System and methods for simultaneous momentum dumping and orbit control

ABSTRACT

The present system and methods enable simultaneous momentum dumping and orbit control of a spacecraft, such as a geostationary satellite. Control equations according to the present system and methods generate accurate station-keeping commands quickly and efficiently, reducing the number of maneuvers needed to maintain station and allowing station-keeping maneuvers to be performed with a single burn. Additional benefits include increased efficiency in propellant usage, and extension of the satellite&#39;s lifespan. The present system and methods also enable tighter orbit control, reduction in transients and number of station-keeping thrusters aboard the satellite. The present methods also eliminate the need for the thrusters to point through the center of mass of the satellite, which in turn reduces the need for dedicated station-keeping thrusters. The present methods also facilitate completely autonomous orbit control and control using Attitude Control Systems (ACS).

BACKGROUND

1. Technical Field

The present disclosure relates to station-keeping for synchronous satellites.

2. Description of Related Art

With reference to FIG. 1, a synchronous satellite 10 orbits the Earth 12 at a rate that matches the Earth's rate of revolution, so that the satellite 10 remains above a fixed point on the Earth 12. FIG. 1 illustrates the satellite 10 at two different points A, B along its orbit path 14. Synchronous satellites are also referred to as geostationary satellites, because they operate within a stationary orbit. Synchronous satellites are used for many applications including weather and communications.

Various forces act on synchronous satellites to perturb their stationary orbits. Examples include the gravitational effects of the sun and the moon, the elliptical shape of the Earth and solar radiation pressure. To counter these forces, synchronous satellites are equipped with propulsion systems that are fired at intervals to maintain station in a desired orbit. For example, the satellite 10 illustrated in FIG. 1 includes a plurality of thrusters 16.

The process of maintaining station, also known as “station-keeping”, requires control of the drift, inclination and eccentricity of the satellite. With reference to FIG. 1, drift is the east-west position of the satellite 10 relative to a sub-satellite point on the Earth 12. Inclination is the north-south position of the satellite 10 relative to the Earth's equator. Eccentricity is the measure of the non-circularity of the satellite orbit 14, or the measure of the variation in the distance between the satellite 10 and the Earth 12 as the satellite 10 orbits the Earth 12. Satellite positioning and orientation is typically controlled from Earth. A control center monitors the satellite's trajectory and issues periodic commands to the satellite to correct orbit perturbations. Typically, orbit control is performed once every two weeks, and momentum dumping is performed every day or every other day.

Current satellites are either spin-stabilized or three-axis stabilized satellites. Spin-stabilized satellites use the gyroscopic effect of the satellite spinning to help maintain the satellite orbit. For certain applications, however, the size of the satellite militates in favor of a three-axis stabilization scheme. Some current three-axis stabilized satellites use separate sets of thrusters to control north-south and east-west motions. The thrusters may burn a chemical propellant or produce an ion discharge, for example, to produce thrust. Alternatively, the thrusters may comprise any apparatus configured to produce a velocity change in the satellite. The north-south thrusters produce the required north-south change in satellite velocity, or ΔV, to control orbit inclination. The east-west thrusters produce the required combined east-west ΔV to control drift and eccentricity. As the cost of satellite propulsion systems is directly related to the number of thrusters required for station keeping, it is advantageous to reduce the number of thrusters required for satellite propulsion and station keeping. Further, propulsion systems have limited lifespans because of the limited supply of fuel onboard the satellite. Thus, it is also advantageous to reduce fuel consumption by onboard thrusters so as to extend the usable life of the satellite.

SUMMARY

The embodiments of the present system and methods for simultaneous momentum dumping and orbit control have several features, no single one of which is solely responsible for their desirable attributes. Without limiting the scope of this system and these methods as expressed by the claims that follow, their more prominent features will now be discussed briefly. After considering this discussion, and particularly after reading the section entitled “Detailed Description”, one will understand how the features of the present embodiments provide advantages, which include a reduction in the number of maneuvers needed to maintain station, increased efficiency in propellant usage, reduction in transients, tighter orbit control, which has the added benefit of reducing the antenna pointing budget, a reduction in the number of station-keeping thrusters needed aboard the satellite, elimination of any need for the thrusters to point through the center of mass of the satellite, thus reducing the need for dedicated station-keeping thrusters, and the potential to enable completely autonomous orbit and ACS control.

One embodiment of the present methods of simultaneous orbit control and momentum dumping in a spacecraft, the spacecraft including a plurality of thrusters, comprises the steps of: generating a set of firing commands for the thrusters from solutions to momentum dumping and inclination control equations; and firing the thrusters according to the firing commands. The momentum dumping and inclination control equations are defined as

$\sqrt{{\Delta \; P_{K_{2}}^{2}} + {\Delta \; P_{H_{2}}^{2}}} = {\Delta \; P_{I}}$ $\lambda_{Inclination} = {a\; \tan \; 2\left( {\frac{\Delta \; P_{H_{2}}}{\Delta \; P_{I}},\frac{\Delta \; P_{K_{2}}}{\Delta \; P_{I}}} \right)}$ ${\Delta \; {\overset{\rightharpoonup}{H}}_{ECI}} = {C_{{Orbit}\mspace{14mu} {to}\mspace{14mu} {ECI}}\Delta \; \overset{\rightharpoonup}{H}}$ ${\Delta \; \overset{\rightharpoonup}{H}} = {\sum\limits_{i}{{{\overset{\rightharpoonup}{r}}_{i} \otimes {\overset{\rightharpoonup}{f}}_{i}}\Delta \; t_{i}}}$ ${{\sum\limits_{i}{f_{i}^{normal}\Delta \; t_{i}}} = {\Delta \; P_{I}}};$

where

Δ{right arrow over (H)}=momentum dumping requirement (vector) in orbit frame

Δ{right arrow over (H)}_(ECI)=momentum dumping requirement (vector) in Earth—Centered Inertial frame

ΔP_(K) ₂ =spacecraft mass×minimum delta velocity required to control mean K₂

ΔP_(H) ₂ =spacecraft mass×minimum delta velocity required to control mean H₂

{right arrow over (R)}_(i)=lever arm (vector) about the c.g. for the i^(th) thruster in spacecraft body frame

{right arrow over (F)}_(i)=thrust vector for the i^(th) thruster in spacecraft body frame

Δt_(i)=on time for the i^(th) thruster

λ_(Inclination)=location of the maneuver

C_(Orbit to ECI)=transformation matrix from orbit to ECI frame,

-   -   rotation matrix about the Z by λ_(Inclination)

C_(Body to Orbit)=transformation matrix from spacecraft body to orbit frame

{right arrow over (r)}_(i)=C_(Body to Orbit) {right arrow over (R)}_(i)

${\overset{\rightharpoonup}{f}}_{i} = {{C_{{Body}\mspace{14mu} {to}\mspace{14mu} {Orbit}}{\overset{\rightharpoonup}{F}}_{i}} = {\begin{bmatrix} f_{i}^{tangential} \\ f_{i}^{radial} \\ f_{i}^{normal} \end{bmatrix}.}}$

Another embodiment of the present methods of simultaneous orbit control and momentum dumping in a spacecraft, the spacecraft including a plurality of thrusters, comprises the steps of: generating a set of firing commands for the thrusters from solutions to momentum dumping and drift control equations; and firing the thrusters according to the firing commands. The momentum dumping and drift control equations are defined as

${\Delta \; \overset{\rightharpoonup}{H}} = {\sum\limits_{i}{{{\overset{\rightharpoonup}{r}}_{i} \otimes {\overset{\rightharpoonup}{f}}_{i}}\Delta \; t_{i}}}$ ${{\sum\limits_{i}{f_{i}^{tangential}\Delta \; t_{i}}} = {\Delta \; P_{Drift}}};$

where

Δ{right arrow over (H)}=momentum dumping requirement (vector) in orbit frame

ΔP_(Drift)=spacecraft mass×minimum delta velocity required to control mean Drift

{right arrow over (R)}_(i)=lever arm (vector) about the c.g. for the i^(th) thruster in spacecraft body frame

{right arrow over (F)}_(i)=thrust vector for the i^(th) thruster in spacecraft body frame

Δt_(i)=on time for the i^(th) thruster

C_(Orbit to ECI)=transformation matrix from orbit to ECI frame

C_(Body to Orbit)=transformation matrix from spacecraft body to orbit frame

{right arrow over (r)}_(i)=C_(Body to Orbit) {right arrow over (R)}_(i)

${\overset{\rightharpoonup}{f}}_{i} = {{C_{{Body}\mspace{14mu} {to}\mspace{11mu} {Orbit}}{\overset{\rightharpoonup}{F}}_{i}} = {\begin{bmatrix} f_{i}^{tangential} \\ f_{i}^{radial} \\ f_{i}^{normal} \end{bmatrix}.}}$

Another embodiment of the present methods simultaneous orbit control and momentum dumping in a spacecraft, the spacecraft including a plurality of thrusters, comprises the steps of: generating a set of firing commands for the thrusters from solutions to momentum dumping/drift and eccentricity control equations; and firing the thrusters according to the firing commands. The momentum dumping/drift and eccentricity control equations are defined as

$P^{tangential} = {\sum\limits_{i}{f_{i}^{tangential}\Delta \; t_{i}}}$ $P^{radial} = {{\sum\limits_{i}{f_{i}^{radial}\Delta \; t_{i}\lambda_{Eccentricity}}} = {\tan^{- 1}\left( \frac{{2P^{tangential}\Delta \; P_{H_{1}}} + {P^{radial}\Delta \; V_{K_{1}}}}{{2P^{tangential}\Delta \; P_{K_{1}}} - {P^{radial}\Delta \; V_{H_{1}}}} \right)}}$ ${{\Delta \; {\overset{\rightharpoonup}{H}}_{ECI}} = {{C_{{Orbit}\mspace{14mu} {to}\mspace{14mu} {ECI}}\Delta \; \overset{\rightharpoonup}{H}{\Delta \; \overset{\rightharpoonup}{H}}} = {{\sum\limits_{i}{{{\overset{\rightharpoonup}{r}}_{i} \otimes {\overset{\rightharpoonup}{f}}_{i}}\Delta \; t_{i}{\sum\limits_{i}{f_{i}^{tangential}\Delta \; t_{i}}}}} = {\Delta \; P_{Drift}}}}};$

where

Δ{right arrow over (H)}=momentum dumping requirement (vector) in orbit frame

Δ{right arrow over (H)}_(ECI)=momentum dumping requirement (vector) in Earth—Centered Inertial frame

ΔP_(K) ₁ =spacecraft mass×minimum delta velocity required to control mean K₁

ΔP_(H) ₁ =spacecraft mass×minimum delta velocity required to control mean H₁

ΔP_(Drift)=spacecraft mass×minimum delta velocity required to control mean Drift

{right arrow over (R)}_(i)=lever arm (vector) about the c.g. for the i^(th) thruster in spacecraft body frame

{right arrow over (F)}_(i)=thrust vector for the i^(th) thruster in spacecraft body frame

Δt_(i)=on time for the i^(th) thruster

λ_(Eccentricity)=location of the maneuver

C_(Orbit to ECI)=transformation matrix from orbit to ECI frame,

-   -   rotation matrix about the Z by λ_(Eccentricity)

C_(Body to Orbit)=transformation matrix from spacecraft body to orbit frame

{right arrow over (r)}_(i)=C_(Body to Orbit) {right arrow over (R)}_(i)

${\overset{\rightharpoonup}{f}}_{i} = {{C_{{Body}\mspace{14mu} {to}\mspace{11mu} {Orbit}}{\overset{\rightharpoonup}{F}}_{i}} = {\begin{bmatrix} f_{i}^{tangential} \\ f_{i}^{radial} \\ f_{i}^{normal} \end{bmatrix}.}}$

Another embodiment of the present methods simultaneous orbit control and momentum dumping in a spacecraft, the spacecraft including a plurality of thrusters, comprises the steps of: generating a set of firing commands for the thrusters from solutions to momentum dumping/drift and eccentricity control equations; and firing the thrusters according to the firing commands. The momentum dumping/drift and eccentricity control equations are defined as

$\mspace{20mu} {{\sum\limits_{{j = 1},2}P_{j}^{tangential}} = {{{\Delta \; {P_{drift}\left( {{2P_{1}^{tangential}\cos \; \lambda_{1}} + {P_{1}^{radial}\sin \; \lambda_{1}}} \right)}} + \left( {{2P_{2}^{tangential}{\cos \left( {\lambda_{1} - {\Delta\lambda}} \right)}} + {P_{2}^{radial}{\sin \left( {\lambda_{1} - {\Delta\lambda}} \right)}}} \right)} = {{{\Delta \; {P_{K_{1}}\left( {{2P_{1}^{tangential}\sin \; \lambda_{1}} - {P_{1}^{radial}\cos \; \lambda_{1}}} \right)}} + \left( {{2P_{2}^{tangential}{\sin \left( {\lambda_{1} - {\Delta\lambda}} \right)}} - {P_{2}^{radial}{\cos \left( {\lambda_{1} - {\Delta\lambda}} \right)}}} \right)} = {{{\Delta \; P_{H_{1}}} - {2P_{1}^{radial}P_{2}^{radial}\sin \; \Delta \; \lambda} - {4P_{1}^{tangential}P_{2}^{radial}\cos \; {\Delta\lambda}} - {8\; P_{1}^{tangential}P_{2}^{tangential}\sin \; {\Delta\lambda}} + {4\; P_{1}^{radial}P_{2}^{tangential}\cos \; \Delta \; \lambda}} = 0}}}}$   λ₂ = λ₁ − Δλ $\mspace{20mu} {{\Delta \; {\overset{\rightharpoonup}{H}}_{ECI}} = {{\Delta \; {\overset{\rightharpoonup}{H}}_{{ECI},1}} + {\Delta \; {\overset{\rightharpoonup}{H}}_{{ECI},2}}}}$ $\mspace{20mu} {{\Delta \; {\overset{\rightharpoonup}{H}}_{{ECI},1}} = {{C_{{Orbit}\mspace{14mu} {to}\mspace{14mu} {ECI}}\left( \lambda_{1} \right)}\Delta \; {\overset{\rightharpoonup}{H}}_{1}}}$ $\mspace{20mu} {{\Delta \; {\overset{\rightharpoonup}{H}}_{{ECI},2}} = {{C_{{Orbit}\mspace{14mu} {to}\mspace{14mu} {ECI}}\left( \lambda_{2} \right)}\Delta \; {\overset{\rightharpoonup}{H}}_{2}}}$ $\mspace{20mu} {P_{j}^{radial} = {\sum\limits_{i}{f_{i,j}^{radial}\Delta \; t_{i,j}}}}$ $\mspace{20mu} {P_{j}^{tangential} = {\sum\limits_{i}{f_{i,j}^{tangential}\Delta \; t_{i,j}}}}$ $\mspace{20mu} {{{\Delta \; {\overset{\rightharpoonup}{H}}_{j}} = {\sum\limits_{i}{{{\overset{\rightharpoonup}{r}}_{i,j} \otimes {\overset{\rightharpoonup}{f}}_{i,j}}\Delta \; t_{i,j}}}};}$

where {right arrow over (r)}_(i,j)=C_(Body to Orbit) {right arrow over (R)}_(i,j)

${\overset{\rightharpoonup}{f}}_{i,j} = {{C_{{Body}\mspace{14mu} {to}\mspace{14mu} {Orbit}}{\overset{\rightharpoonup}{F}}_{i,j}} = \begin{bmatrix} f_{i,j}^{tangential} \\ f_{i,j}^{radial} \\ f_{i,j}^{normal} \end{bmatrix}}$ j = 1, 2 i = index  for  the  i^(th)  thruster.

One embodiment of the present system for simultaneous orbit control and momentum dumping of a spacecraft comprises a spacecraft including a plurality of thrusters, and means for generating a set of firing commands for the thrusters from solutions to momentum dumping and inclination control equations. The momentum dumping and inclination control equations are defined as

$\sqrt{{\Delta \; P_{K_{2}}^{2}} + {\Delta \; P_{H_{2}}^{2}}} = {\Delta \; P_{I}}$ $\lambda_{Inclination} = {a\; \tan \; 2\left( {\frac{\Delta \; P_{H_{2}}}{\Delta \; P_{I}},\frac{\Delta \; P_{K_{2}}}{\Delta \; P_{I}}} \right)}$ ${\Delta \; {\overset{\rightharpoonup}{H}}_{ECI}} = {C_{{Orbit}\mspace{14mu} {to}\mspace{14mu} {ECI}}\Delta \; \overset{\rightharpoonup}{H}}$ ${\Delta \; \overset{\rightharpoonup}{H}} = {\sum\limits_{i}{{{\overset{\rightharpoonup}{r}}_{i} \otimes {\overset{\rightharpoonup}{f}}_{i}}\Delta \; t_{i}}}$ ${{\sum\limits_{i}{f_{i}^{normal}\Delta \; t_{i}}} = {\Delta \; P_{I}}};$

where

Δ{right arrow over (H)}=momentum dumping requirement (vector) in orbit frame

Δ{right arrow over (H)}_(ECI)=momentum dumping requirement (vector) in Earth—Centered Inertial frame

ΔP_(K) ₂ =spacecraft mass×minimum delta velocity required to control mean K₂

ΔP_(H) ₂ =spacecraft mass×minimum delta velocity required to control mean H₂

{right arrow over (R)}_(i)=lever arm (vector) about the c.g. for the i^(th) thruster in spacecraft body frame {right arrow over (F)}_(i)=thrust vector for the i^(th) thruster in spacecraft body frame

Δt_(i)=on time for the i^(th) thruster

λ_(Inclination)=location of the maneuver

C_(Orbit to ECI)=transformation matrix from orbit to ECI frame,

-   -   rotation matrix about the Z by λ_(Inclination)

C_(Body to Orbit)=transformation matrix from spacecraft body to orbit frame

{right arrow over (r)}_(i)=C_(Body to Orbit) {right arrow over (R)}_(i)

${\overset{\rightharpoonup}{f}}_{i} = {{C_{{Body}\mspace{14mu} {to}\mspace{11mu} {Orbit}}{\overset{\rightharpoonup}{F}}_{i}} = {\begin{bmatrix} f_{i}^{tangential} \\ f_{i}^{radial} \\ f_{i}^{normal} \end{bmatrix}.}}$

Another embodiment of the present system for simultaneous orbit control and momentum dumping of a spacecraft comprises a spacecraft configured to orbit Earth in a geostationary orbit, and further configured to autonomously control a position of the spacecraft relative to a fixed point on Earth. The spacecraft further comprises a spacecraft body and a plurality of thrusters associated with the spacecraft body. The spacecraft generates a set of firing commands for the thrusters from solutions to momentum dumping and inclination control equations, and the spacecraft fires the thrusters according to the firing commands. The momentum dumping and inclination control equations are defined as

$\sqrt{{\Delta \; P_{K_{2}}^{2}} + {\Delta \; P_{H_{2}}^{2}}} = {\Delta \; P_{I}}$ $\lambda_{Inclination} = {a\; \tan \; 2\left( {\frac{\Delta \; P_{H_{2}}}{\Delta \; P_{I}},\frac{\Delta \; P_{K_{2}}}{\Delta \; P_{I}}} \right)}$ ${\Delta \; {\overset{\rightharpoonup}{H}}_{ECI}} = {C_{{Orbit}\mspace{14mu} {to}\mspace{14mu} {ECI}}\Delta \; \overset{\rightharpoonup}{H}}$ ${\Delta \; \overset{\rightharpoonup}{H}} = {\sum\limits_{i}{{{\overset{\rightharpoonup}{r}}_{i} \otimes {\overset{\rightharpoonup}{f}}_{i}}\Delta \; t_{i}}}$ ${{\sum\limits_{i}{f_{i}^{normal}\Delta \; t_{i}}} = {\Delta \; P_{I}}};$

where

Δ{right arrow over (H)}=momentum dumping requirement (vector) in orbit frame

Δ{right arrow over (H)}_(ECI)=momentum dumping requirement (vector) in Earth—Centered Inertial frame

ΔP_(K) ₂ =spacecraft mass×minimum delta velocity required to control mean K₂

ΔP_(H) ₂ =spacecraft mass×minimum delta velocity required to control mean H₂

{right arrow over (R)}_(i)=lever arm (vector) about the c.g. for the i^(th) thruster in spacecraft body frame

{right arrow over (F)}_(i)=thrust vector for the i^(th) thruster in spacecraft body frame

Δt_(i)=on time for the i^(th) thruster

λ_(Inclination)=location of the maneuver

C_(Orbit to ECI)=transformation matrix from orbit to ECI frame,

-   -   rotation matrix about the Z by λ_(Inclination)

C_(Body to Orbit)=transformation matrix from spacecraft body to orbit frame

{right arrow over (r)}_(i)=C_(Body to Orbit) {right arrow over (R)}_(i)

${\overset{\rightharpoonup}{f}}_{i} = {{C_{{Body}\mspace{14mu} {to}\mspace{14mu} {Orbit}}{\overset{\rightharpoonup}{F}}_{i}} = {\begin{bmatrix} f_{i}^{tangential} \\ f_{i}^{radial} \\ f_{i}^{normal} \end{bmatrix}.}}$

The features, functions, and advantages of the present embodiments can be achieved independently in various embodiments or may be combined in yet other embodiments.

BRIEF DESCRIPTION OF THE DRAWINGS

The embodiments of the present system and methods for simultaneous momentum dumping and orbit control will now be discussed in detail with an emphasis on highlighting the advantageous features. These embodiments depict the novel and non-obvious system and methods shown in the accompanying drawings, which are for illustrative purposes only. These drawings include the following figures, in which like numerals indicate like parts:

FIG. 1 is a front perspective view of a geostationary satellite orbiting the Earth.

DETAILED DESCRIPTION

In describing the present embodiments, the following symbols will be used:

Eccentricity(e) vector: Σ=Ω+tan⁻¹(tan(ω)cos(i)) h₁=e sin (Σ) k₁=e cos (Σ) Inclination(i) vector: h₂=sin (i) sin Ω. k₂=sin (i) cos Ω. Ω=right ascension of ascending node ω=argument of perigee I=i=inclination of the orbit

${{mean}\mspace{14mu} {drift}\mspace{14mu} {rate}} = \left\lbrack {{\frac{2\pi}{{Period}_{Nominal}}\sqrt{\frac{a^{3}}{\mu}}} - 1} \right\rbrack$

a=semi−major axis Period_(Normal)=nominal orbital period of the desired orbit V_(synchronous)=orbital velocity at geosynchronous orbit R_(synchronous)=distance from center of the Earth at geosynchronous orbit ΔV_(i)=magnitude of the delta velocity for i^(th) maneuver t_(i)=direction cosine of ΔV_(i) along orbit tangential direction n_(i)=direction cosine of ΔV_(i) along orbit normal direction r_(i)=direction cosine of ΔV_(i) along orbit radial direction λ_(i)=applied delta velocity right ascension ΔV_(ion)=minimum delta velocity required for change of argument of latitude (*mean longitude) ΔV_(drift)=minimum delta velocity required to control mean semi-major axis (*longitudinal drift) ΔV_(K) ₁ =minimum delta velocity required to control mean K₁ ΔV_(H) ₁ =minimum delta velocity required to control mean H₁ ΔV_(K) ₂ =minimum delta velocity required to control mean K₂ ΔV_(H) ₂ =minimum delta velocity required to control mean H₂ *For geosynchronous orbit To control orbit, the size(s) (ΔV) and location(s) (X) of the maneuver(s) that can correct the orbit must be found. The basic control equations for drift and eccentricity control are:

${\sum\limits_{{i = 1},2}^{\;}\; {\Delta \; V_{i}t_{i}}} = {\Delta \; V_{drift}}$ ${\sum\limits_{{i = 1},2}^{\;}\; {\Delta \; {V_{i}\left( {{2t_{i}\cos \; \lambda_{i}} + {r_{i}\sin \; \lambda_{i}}} \right)}}} = {\Delta \; V_{K_{1}}}$ ${\sum\limits_{{i = 1},2}^{\;}\; {\Delta \; {V_{i}\left( {{2t_{i}\sin \; \lambda_{i}} - {r_{i}\cos \; \lambda_{i}}} \right)}}} = {\Delta \; V_{H_{1}}}$

And the basic control equations for inclination control are:

ΔV₃n₃ cos λ₃=ΔV_(K) ₂

ΔV₃n₃ sin λ₃=ΔV_(H) ₂

Under some circumstances, a set of three burns may be used to control the longitudinal drift rate, eccentricity [K₁ H₁], and inclination [K₂ H₂] for a satellite in near geo-stationary orbit. From the equations and symbols above, then:

${\sum\limits_{{i = 1},3}^{\;}\; {\Delta \; V_{i}t_{i}}} = {\Delta \; V_{lon}}$ ${\sum\limits_{{i = 1},3}^{\;}\; {\Delta \; V_{i}t_{i}}} = {\Delta \; V_{drift}}$ ${\sum\limits_{{i = 1},3}^{\;}\; {\Delta \; {V_{i}\left( {{2t_{i}\cos \; \lambda_{i}} + {r_{i}\sin \; \lambda_{i}}} \right)}}} = {\Delta \; V_{K_{1}}}$ ${\sum\limits_{{i = 1},3}^{\;}\; {\Delta \; {V_{i}\left( {{2t_{i}\sin \; \lambda_{i}} - {r_{i}\cos \; \lambda_{i}}} \right)}}} = {\Delta \; V_{H_{1}}}$ ${\sum\limits_{{i = 1},3}^{\;}\; {\Delta \; V_{i}n_{i}\cos \; \lambda_{i}}} = {\Delta \; V_{K_{2}}}$ ${\sum\limits_{{i = 1},3}^{\;}\; {\Delta \; V_{i}n_{i}\sin \; \lambda_{i}}} = {\Delta \; V_{H_{2}}}$

Under some circumstances, however, the longitude equation above may not be used. For example, after orbit initialization the satellite is at the nominal longitude location. Then only the longitudinal drift may need to be corrected in order to keep the longitude error to within a desired range, such as, for example ±0.05°. Therefore, the remaining five equations form the basis for the maneuver calculation. In some situations these equations cannot be solved analytically. However, careful choices regarding, for example, thruster locations and orientations and satellite configurations can simplify their solutions.

Propellant consumption is sometimes the primary concern for chemical propulsion systems. Therefore, station-keeping thrusters may be configured specifically either for north/south (inclination control) or east/west (drift and eccentricity control) maneuvers with minimal unwanted components. Under these conditions the set of equations above becomes:

${\sum\limits_{{i = 1},2}^{\;}\; {\Delta \; V_{i}t_{i}}} = {\Delta \; V_{drift}}$ ${\sum\limits_{{i = 1},2}^{\;}\; {\Delta \; {V_{i}\left( {{2t_{i}\cos \; \lambda_{i}} + {r_{i}\sin \; \lambda_{i}}} \right)}}} = {\Delta \; V_{K_{1}}}$ ${\sum\limits_{{i = 1},2}^{\;}\; {\Delta \; {V_{i}\left( {{2t_{i}\sin \; \lambda_{i}} - {r_{i}\cos \; \lambda_{i}}} \right)}}} = {\Delta \; V_{H_{1}}}$ Δ V₃n₃cos  λ₃ = Δ V_(K₂) Δ V₃n₃sin  λ₃ = Δ V_(H₂)

with the first three equations above controlling drift and eccentricity and the last two equations controlling inclination.

For maneuver planning, the size(s) (ΔV) and location(s) (X) of the burn(s) that can correct the orbit according to the selected control strategy must be found. For a given ΔV_(drift) and [ΔV_(K1) ΔV_(H1)], one can solve for the two sets of ΔV's and λ's analytically by reformulating the equations for drift and eccentricity control:

$\mspace{79mu} {{\sum\limits_{{i = 1},2}^{\;}\; {\Delta \; V_{i}t_{i}}} = {\Delta \; V_{drift}}}$ Δ V₁(2 t₁cos  λ₁ + r₁sin  λ₁) + Δ V₂(2 t₂cos  (λ₁ − Δλ) + r₂sin (λ₁ − Δλ)) = Δ V_(K₁) Δ V₁(2 t₁sin  λ₁ − r₁cos  λ₁) + Δ V₂(2 t₂sin  (λ₁ − Δλ) + r₂cos (λ₁ − Δλ)) = Δ V_(H₁) − 2Δ V₁r₁Δ V₂r₂sin  Δλ − 4Δ V₁t₁Δ V₂r₂cos  Δλ − 8Δ V₁t₁Δ V₂t₂sin  Δλ + 4Δ V₁r₁Δ V₂t₂cos  Δλ = 0

where λ₂=λ₁−Δλ

In the equations above there are four possible solutions for ΔV₁, ΔV₂, λ₁ and Δλ:

${\Delta \; V_{1}} = \begin{Bmatrix} {\sqrt{B}\begin{matrix} {\begin{pmatrix} {{16\frac{\Delta \; V_{drift}t_{1}^{2}t_{2}^{2}}{\sqrt{AB}}} + {4\frac{\Delta \; V_{drift}t_{1}^{2}r_{2}^{2}}{\sqrt{AB}}} +} \\ {\frac{\Delta \; V_{drift}r_{1}^{2}r_{2}^{2}}{\sqrt{AB}} + {4\frac{\Delta \; V_{drift}t_{2}^{2}r_{1}^{2}}{\sqrt{AB}}} - t_{2}} \end{pmatrix}/} \\ {\left( {{4t_{2}^{2}} + r_{1}^{2}} \right)\left( {{4\frac{t_{2}^{2}t_{1}}{\sqrt{A}}} + \frac{t_{1}r_{2}^{2}}{\sqrt{A}} - t_{2}} \right)} \end{matrix}} \\ {\sqrt{B}\begin{matrix} {\begin{pmatrix} {{16\frac{\Delta \; V_{drift}t_{1}^{2}t_{2}^{2}}{\sqrt{AB}}} + {4\frac{\Delta \; V_{drift}t_{1}^{2}r_{2}^{2}}{\sqrt{AB}}} +} \\ {\frac{\Delta \; V_{drift}r_{1}^{2}r_{2}^{2}}{\sqrt{AB}} + {4\frac{\Delta \; V_{drift}t_{2}^{2}r_{1}^{2}}{\sqrt{AB}}} + t_{2}} \end{pmatrix}/} \\ {\left( {{4t_{2}^{2}} + r_{1}^{2}} \right)\left( {{4\frac{t_{2}^{2}t_{1}}{\sqrt{A}}} + \frac{t_{1}r_{2}^{2}}{\sqrt{A}} - t_{2}} \right)} \end{matrix}} \\ {\sqrt{B}\begin{matrix} {\begin{pmatrix} {{16\frac{\Delta \; V_{drift}t_{1}^{2}t_{2}^{2}}{\sqrt{AB}}} + {4\frac{\Delta \; V_{drift}t_{1}^{2}r_{2}^{2}}{\sqrt{AB}}} +} \\ {\frac{\Delta \; V_{drift}r_{1}^{2}r_{2}^{2}}{\sqrt{AB}} + {4\frac{\Delta \; V_{drift}t_{2}^{2}r_{1}^{2}}{\sqrt{AB}}} + t_{2}} \end{pmatrix}/} \\ {\left( {{4t_{2}^{2}} + r_{1}^{2}} \right)\left( {{4\frac{t_{2}^{2}t_{1}}{\sqrt{A}}} + \frac{t_{1}r_{2}^{2}}{\sqrt{A}} + t_{2}} \right)} \end{matrix}} \\ {\sqrt{B}\begin{matrix} {\begin{pmatrix} {{16\frac{\Delta \; V_{drift}t_{1}^{2}t_{2}^{2}}{\sqrt{AB}}} + {4\frac{\Delta \; V_{drift}t_{1}^{2}r_{2}^{2}}{\sqrt{AB}}} +} \\ {\frac{\Delta \; V_{drift}r_{1}^{2}r_{2}^{2}}{\sqrt{AB}} + {4\frac{\Delta \; V_{drift}t_{2}^{2}r_{1}^{2}}{\sqrt{AB}}} - t_{2}} \end{pmatrix}/} \\ {\left( {{4t_{2}^{2}} + r_{1}^{2}} \right)\left( {{4\frac{t_{2}^{2}t_{1}}{\sqrt{A}}} + \frac{t_{1}r_{2}^{2}}{\sqrt{A}} + t_{2}} \right)} \end{matrix}} \end{Bmatrix}$ A = 4t₁²r₂² + 4r₁²t₂² + r₁²r₂² + 16t₁²t₂² B = 4t₁²Δ V_(H₁)² + 4₁²Δ V_(K₁)² + r₁²Δ V_(K₁)² + r₁²Δ V_(H₁)² ${\Delta \; V_{2}} = \begin{Bmatrix} \begin{matrix} \begin{matrix} \begin{matrix} {{- \Delta}\; {{V_{drift}\left( {{4\Delta \; V_{drift}t_{1}^{2}} + r_{1}^{2} + {t_{1}\sqrt{B}}} \right)}/}} \\ {\left( {{4t_{2}^{2}} + r_{1}^{2}} \right)\left( {{4\frac{t_{2}^{2}t_{1}}{\sqrt{A}}} + \frac{t_{1}r_{2}^{2}}{\sqrt{A}} - t_{2}} \right)} \end{matrix} \\ \begin{matrix} {{- \Delta}\; {{V_{drift}\left( {{4\Delta \; V_{drift}t_{1}^{2}} + r_{1}^{2} + {t_{1}\sqrt{B}}} \right)}/}} \\ {\left( {{4t_{2}^{2}} + r_{1}^{2}} \right)\left( {{4\frac{t_{2}^{2}t_{1}}{\sqrt{A}}} + \frac{t_{1}r_{2}^{2}}{\sqrt{A}} - t_{2}} \right)} \end{matrix} \end{matrix} \\ \begin{matrix} {\Delta \; {{V_{drift}\left( {{4\Delta \; V_{drift}t_{1}^{2}} + r_{1}^{2} - {t_{1}\sqrt{B}}} \right)}/}} \\ {\left( {{4t_{2}^{2}} + r_{1}^{2}} \right)\left( {{4\frac{t_{2}^{2}t_{1}}{\sqrt{A}}} + \frac{t_{1}r_{2}^{2}}{\sqrt{A}} + t_{2}} \right)} \end{matrix} \end{matrix} \\ \begin{matrix} {\Delta \; {{V_{drift}\left( {{4\Delta \; V_{drift}t_{1}^{2}} + r_{1}^{2} + {t_{1}\sqrt{B}}} \right)}/}} \\ {\left( {{4t_{2}^{2}} + r_{1}^{2}} \right)\left( {{4\frac{t_{2}^{2}t_{1}}{\sqrt{A}}} + \frac{t_{1}r_{2}^{2}}{\sqrt{A}} + t_{2}} \right)} \end{matrix} \end{Bmatrix}$ A = 4t₁²r₂² + 4r₁²t₂² + r₁²r₂² + 16t₁²t₂² B = 4t₁²Δ V_(H₁)² + 4₁²Δ V_(K₁)² + r₁²Δ V_(K₁)² + r₁²Δ V_(H₁)² $\lambda_{1} = \begin{Bmatrix} \begin{matrix} \begin{matrix} {a\; \tan \; 2\left( {\frac{{r_{1}\Delta \; V_{K_{1}}} + {2t_{1}\Delta \; V_{H_{1}}}}{\sqrt{B}},\frac{{2t_{1}\Delta \; V_{K_{1}}} - {r_{1}\Delta \; V_{H_{1}}}}{\sqrt{B}}} \right)} \\ {a\; \tan \; 2\left( {{- \frac{{r_{1}\Delta \; V_{K_{1}}} + {2t_{1}\Delta \; V_{H_{1}}}}{\sqrt{B}}},\frac{{2t_{1}\Delta \; V_{K_{1}}} - {r_{1}\Delta \; V_{H_{1}}}}{\sqrt{B}}} \right)} \end{matrix} \\ {a\; \tan \; 2\left( {\frac{{r_{1}\Delta \; V_{K_{1}}} + {2t_{1}\Delta \; V_{H_{1}}}}{\sqrt{B}},\frac{{2t_{1}\Delta \; V_{K_{1}}} - {r_{1}\Delta \; V_{H_{1}}}}{\sqrt{B}}} \right)} \end{matrix} \\ {a\; \tan \; 2\left( {{- \frac{{r_{1}\Delta \; V_{K_{1}}} + {2t_{1}\Delta \; V_{H_{1}}}}{\sqrt{B}}},\frac{{2t_{1}\Delta \; V_{K_{1}}} - {r_{1}\Delta \; V_{H_{1}}}}{\sqrt{B}}} \right)} \end{Bmatrix}$ ${\Delta\lambda} = \begin{Bmatrix} \begin{matrix} \begin{matrix} {a\; \tan \; 2\left( {\frac{2\left( {{t_{2}r_{1}} - {t_{1}r_{2}}} \right)}{\sqrt{A}},\frac{{r_{1}r_{2}} + {4t_{1}t_{2}}}{\sqrt{A}}} \right)} \\ {a\; \tan \; 2\left( {\frac{2\left( {{t_{2}r_{1}} - {t_{1}r_{2}}} \right)}{\sqrt{A}},\frac{{r_{1}r_{2}} + {4t_{1}t_{2}}}{\sqrt{A}}} \right)} \end{matrix} \\ {a\; \tan \; 2\left( {{- \frac{2\left( {{t_{2}r_{1}} - {t_{1}r_{2}}} \right)}{\sqrt{A}}},\frac{{r_{1}r_{2}} + {4t_{1}t_{2}}}{\sqrt{A}}} \right)} \end{matrix} \\ {a\; \tan \; 2\left( {{- \frac{2\left( {{t_{2}r_{1}} - {t_{1}r_{2}}} \right)}{\sqrt{A}}},\frac{{r_{1}r_{2}} + {4t_{1}t_{2}}}{\sqrt{A}}} \right)} \end{Bmatrix}$

The solution to the above equations that provides the minimum ΔV₁ and ΔV₂ is the most advantageous choice, since smaller velocity changes generally consume less fuel than larger velocity changes, and since smaller velocity changes have less potential to create unwanted disturbances in the satellite's orbit as compared to larger velocity changes. However, the solution becomes invalid if either ΔV₁ or ΔV₂ is less than zero, which occurs when the magnitude of ΔV_(drift) approaches the magnitude of [ΔN_(K1) ΔV_(H1)]. In these situations the formulation for one maneuver can be used, and one set of ΔV and λ control both the drift and eccentricity:

${\Delta \; V_{1}} = \frac{\Delta \; V_{drift}}{t_{1}}$ $\lambda_{1} = {\tan^{- 1}\left( \frac{{\Delta \; V_{1}2t_{1}\Delta \; V_{H_{1}}} + {\Delta \; V_{1}r_{1}\Delta \; V_{K_{1}}}}{{\Delta \; V_{1}2t_{1}\Delta \; V_{K_{1}}} - {\Delta \; V_{1}r_{1}\Delta \; V_{H_{1}}}} \right)}$

According to the equations above, the size of the burn is dictated by the drift correction while the location of the burn is determined by the direction of the eccentricity correction [ΔV_(K1) ΔV_(H1)] and the in-plane components of the thrust vector [t₁ r₁]. Since ΔV_(drift) does not necessarily have the same magnitude as [ΔV_(K1) ΔV_(H1)], the one maneuver solution may result in either under correction (undershoot) or over correction (overshoot) of the eccentricity perturbation. In such cases, the difference can be corrected in the next control cycle. For a given inclination correction [ΔV_(K2) ΔV_(H2)], the solutions for ΔV and λ are very simple:

${\Delta \; V_{I}} = \sqrt{{\Delta \; V_{H_{2}}^{2}} + {\Delta \; V_{K_{2}}^{2}}}$ ${\Delta \; V_{3}} = \frac{\Delta \; V_{I}}{n_{3}}$ $\lambda_{3} = {a\; \tan \; 2\left( {\frac{\Delta \; V_{H_{2}}}{\Delta \; V_{I}},\frac{\Delta \; V_{K_{2}}}{\Delta \; V_{I}}} \right)}$

According to the present embodiments, it is possible to perform simultaneous momentum dumping and orbit control. Benefits achieved by the present embodiments include a reduction in the number of maneuvers needed to maintain station, increased efficiency in propellant usage, reduction in transients, tighter orbit control, which has the added benefit of reducing the antenna pointing budget, a reduction in the number of station-keeping thrusters needed aboard the satellite, elimination of any need for the thrusters to point through the center of mass of the satellite, thus reducing the need for dedicated station-keeping thrusters, and the potential to enable completely autonomous orbit and ACS control.

In the present embodiments, since the equations for orbit control are in the orbit frame, the momentum dumping requirement is computed in the same frame:

Δ{right arrow over (H)}=momentum dumping requirement (vector) in orbit frame

Δ{right arrow over (H)}_(ECI)=momentum dumping requirement (vector) in Earth—Centered Inertial frame

{right arrow over (R)}_(i)=lever arm (vector) about the c.g. for the i^(th) thruster in spacecraft body frame

{right arrow over (F)}_(i)=thrust vector for the i^(th) thruster in spacecraft body frame

Δt_(i)=on time for the i^(th) thruster

C_(Orbit to ECI)=transformation matrix from orbit to ECI frame,

C_(Body to Orbit)=transformation matrix from spacecraft body to orbit frame

{right arrow over (r)}_(i)=C_(Body to Orbit) {right arrow over (R)}_(i)

{right arrow over (f)}_(i)=C_(Body to Orbit) {right arrow over (F)}

${\Delta \; \overset{\rightharpoonup}{H}} = {\sum\limits_{i}\; {{{\overset{\rightharpoonup}{r}}_{i} \otimes {\overset{\rightharpoonup}{f}}_{i}}\Delta \; t_{i}}}$

Δ{right arrow over (H)}_(ECI)=C_(Orbit to ECI)Δ{right arrow over (H)}

Using the equation for impulse,

{right arrow over (P)}(impulse)={right arrow over (f)}(thrust)Δt(ontime)=M (spacecraft_mass)Δ{right arrow over (V)}(delta_velocity), the equations for momentum and orbit control can be reformulated into more convenient forms by multiplying the orbit control equations by the spacecraft mass, which changes very little for small burns:

$\mspace{20mu} {{M{\sum\limits_{i}^{\;}\; {\Delta \; V_{i}t_{i}}}} = {{{M\; \Delta \; V_{drift}}{\sum\limits_{i}^{\;}\; {f_{i}^{tangential}\Delta \; t_{i}}}} = {\Delta \; P_{drift}}}}$ ${M{\sum\limits_{i}^{\;}\; {\Delta \; {V_{i}\left( {{2t_{i}\cos \; \lambda_{i}} + {r_{i}\sin \; \lambda_{i}}} \right)}}}} = {\left. {M\; \Delta \; V_{K_{1}}}\rightarrow{\sum\limits_{i}^{\;}\; {\begin{pmatrix} {{2f_{i}^{tangential}\cos \; \lambda_{i}} +} \\ {f_{i}^{radial}\sin \; \lambda_{i}} \end{pmatrix}{\Delta t}_{i}}} \right. = {\Delta \; P_{K_{1}}}}$ ${M{\sum\limits_{i}^{\;}\; {\Delta \; {V_{i}\left( {{2t_{i}\sin \; \lambda_{i}} + {r_{i}\cos \; \lambda_{i}}} \right)}}}} = {\left. {M\; \Delta \; V_{H_{1}}}\rightarrow{\sum\limits_{i}^{\;}\; {\begin{pmatrix} {{2f_{i}^{tangential}\sin \; \lambda_{i}} +} \\ {f_{i}^{radial}\cos \; \lambda_{i}} \end{pmatrix}{\Delta t}_{i}}} \right.\; = {\Delta \; P_{H_{1}}}}$ $\mspace{79mu} {{M{\sum\limits_{i}^{\;}\; {\Delta \; V_{i}n_{i}\cos \; \lambda_{i}}}} = {\left. {M\; \Delta \; V_{K_{2}}}\rightarrow{\sum\limits_{i}^{\;}\; {\left( {f_{i}^{normal}\cos \; \lambda_{i}} \right)\Delta \; t_{i}}} \right. = {\Delta \; P_{K_{2}}}}}$ $\mspace{20mu} {{M{\sum\limits_{i}^{\;}\; {\Delta \; V_{i}n_{i}\sin \; \lambda_{i}}}} = {\left. {M\; \Delta \; V_{H_{2}}}\rightarrow{\sum\limits_{i}^{\;}\; {\left( {f_{i}^{normal}\sin \; \lambda_{i}} \right)\Delta \; t_{i}}} \right. = {\Delta \; P_{H_{2}}}}}$ $\mspace{20mu} {{\Delta \overset{\rightharpoonup}{H}} = {\left. {\sum\limits_{i}^{\;}\; {{{\overset{\rightharpoonup}{r}}_{i} \otimes {\overset{\rightharpoonup}{f}}_{i}}\Delta \; t_{i}}}\rightarrow{\Delta \; \overset{\rightharpoonup}{H}} \right. = {\sum\limits_{i}^{\;}\; {{\overset{\rightharpoonup}{r}}_{i} \otimes {\overset{\rightharpoonup}{P}}_{i}}}}}$

There are eight equations above, five for the orbit control and three for the momentum dump. Accordingly, the equations require eight unknowns for their solutions. However, since the orientation of ΔH (the momentum vector in the orbit frame) varies with orbital position of the spacecraft, closed form solutions to the eight equations above can be found by coupling the momentum dumping with orbit control in specific directions. For example, coupling the momentum dumping with drift control yields the following simple algebraic equations:

${\sum\limits_{i}^{\;}\; {f_{i}^{tangential}\Delta \; t_{i}}} = {\Delta \; P_{drift}}$ ${\Delta \; \overset{\rightharpoonup}{H}} = {\sum\limits_{i}^{\;}\; {{\overset{\rightharpoonup}{r}}_{i} \otimes {\overset{\rightharpoonup}{P}}_{i}}}$

And coupling the momentum dumping with inclination control yields the following equations:

$\sqrt{{\Delta \; P_{H_{2}}^{2}} + {\Delta \; P_{K_{2}}^{2}}} = {\Delta \; P_{I}}$ ${\sum\limits_{i}^{\;}\; {f_{i}^{normal}\Delta \; t_{i}}} = {\Delta \; P_{I}}$ ${\Delta \; \overset{\rightharpoonup}{H}} = {\sum\limits_{i}^{\;}\; {{\overset{\rightharpoonup}{r}}_{i} \otimes {\overset{\rightharpoonup}{P}}_{i}}}$

Either set of equations above requires just four unknowns for their general solutions. For a satellite with fixed thrusters, the unknown can be chosen as the on time of the thrusters. Therefore, the momentum dumping and the selected orbit control can advantageously be accomplished by firing thrusters without the need to mount the thrusters on gimbaled platforms. The momentum dump can be performed in conjunction with drift control, or in conjunction with inclination control, or a combination of both.

By solving for the location of the maneuver, the complete solution for the momentum dumping and inclination control can easily be obtained from the following equations:

$\sqrt{{\Delta \; P_{K_{2}}^{2}} + {\Delta \; P_{H_{2}}^{2}}} = {\Delta \; P_{I}}$ $\lambda_{Inclination} = {a\; \tan \; 2\left( {\frac{\Delta \; P_{H_{2}}}{\Delta \; P_{I}},\frac{\Delta \; P_{K_{2}}}{\Delta \; P_{I}}} \right)}$ ${\Delta \; \overset{\rightharpoonup}{H}} = {C_{{Orbit}\mspace{14mu} {to}\mspace{14mu} {ECI}}^{- 1}\Delta \; {\overset{\rightharpoonup}{H}}_{ECI}}$ ${\sum\limits_{i}^{\;}\; {{{\overset{\rightharpoonup}{r}}_{i} \otimes {\overset{\rightharpoonup}{f}}_{i}}\Delta \; t_{i}}} = {\Delta \; \overset{\rightharpoonup}{H}}$ ${\sum\limits_{i}^{\;}\; {f_{i}^{normal}\Delta \; t_{i}}} = {\Delta \; P_{1}}$

where

Δ{right arrow over (H)}=momentum dumping requirement (vector) in orbit frame

Δ{right arrow over (H)}_(ECI)=momentum dumping requirement (vector) in Earth—Centered Inertial frame

ΔP_(K) ₂ =spacecraft mass×minimum delta velocity required to control mean K₂

ΔP_(H) ₂ =spacecraft mass×minimum delta velocity required to control mean H₂

{right arrow over (R)}_(i)=lever arm (vector) about the c.g. for the i^(th) thruster in spacecraft body frame

{right arrow over (F)}_(i)=thrust vector for the i^(th) thruster in spacecraft body frame

Δt_(i)=on time for the i^(th) thruster

λ_(Inclination)=location of the maneuver

C_(Orbit to ECI)=transformation matrix from orbit to ECI frame,

-   -   rotation matrix about the Z by λ_(Inclination)

C_(Body to Orbit)=transformation matrix from spacecraft body to orbit frame

{right arrow over (r)}_(i)=C_(Body to Orbit) {right arrow over (R)}_(i)

${\overset{\rightharpoonup}{f}}_{i} = {{C_{{Body}\mspace{14mu} {to}\mspace{14mu} {Orbit}}{\overset{\rightharpoonup}{F}}_{i}} = \begin{bmatrix} f_{i}^{tangential} \\ f_{i}^{radial} \\ f_{i}^{normal} \end{bmatrix}}$

Since the maneuver to control the drift is independent of location, the complete solution for the momentum dumping and drift control can be obtained from the following algebraic equations:

${\sum\limits_{i}^{\;}\; {f_{i}^{tangential}\Delta \; t_{i}}} = {\Delta \; P_{Drift}}$ ${\sum\limits_{i}^{\;}\; {{{\overset{\rightharpoonup}{r}}_{i} \otimes {\overset{\rightharpoonup}{f}}_{i}}\Delta \; t_{i}}} = {\Delta \; \overset{\rightharpoonup}{H}}$

where

Δ{right arrow over (H)}=momentum dumping requirement (vector) in orbit frame

ΔP_(Drift)=spacecraft mass×minimum delta velocity required to control mean Drift

{right arrow over (R)}_(i)=lever arm (vector) about the c.g. for the i^(th) thruster in spacecraft body frame

{right arrow over (F)}_(i)=thrust vector for the i^(th) thruster in spacecraft body frame

Δt_(i)=on time for the i^(th) thruster

C_(Orbit to ECI)=transformation matrix from orbit to ECI frame

C_(Body to Orbit)=transformation matrix from spacecraft body to orbit frame

{right arrow over (r)}_(i)=C_(Body to Orbit) {right arrow over (R)}_(i)

${\overset{\rightharpoonup}{f}}_{i} = {{C_{{Body}\mspace{14mu} {to}\mspace{14mu} {Orbit}}{\overset{\rightharpoonup}{F}}_{i}} = \begin{bmatrix} f_{i}^{tangential} \\ f_{i}^{radial} \\ f_{i}^{normal} \end{bmatrix}}$

By placing the drift maneuvers in the locations determined by the drift and eccentricity control equations, the momentum dumping can be performed in conjunction with the eccentricity control. For one maneuver drift and eccentricity control, λ_(Eccentricity) can be found by simple iteration (or root searching method) of the following equations:

$P^{radial} = {\sum\limits_{i}\; {f_{i}^{radial}\Delta \; t_{i}}}$ $\lambda_{Eccentricity} = {\tan^{- 1}\left( \frac{{2\Delta \; P_{Drift}\Delta \; P_{H_{1}}} + {P^{radial}\Delta \; P_{K_{1}}}}{{2\Delta \; P_{Drift}\Delta \; P_{K_{1}}} - {P^{radial}\Delta \; P_{H_{1}}}} \right)}$ ${\Delta \; \overset{\rightharpoonup}{H}} = {C_{{Orbit}\mspace{14mu} {to}\mspace{14mu} {ECI}}^{- 1}\Delta \; {\overset{\rightharpoonup}{H}}_{ECI}}$ ${\sum\limits_{i}{{{\overset{\rightharpoonup}{r}}_{i} \otimes {\overset{\rightharpoonup}{f}}_{i}}\Delta \; t_{i}}} = {\Delta \overset{\rightharpoonup}{H}}$ ${\sum\limits_{i}\; {f_{i}^{tangential}\Delta \; t_{i}}} = {\Delta \; P_{Drift}}$

where

Δ{right arrow over (H)}=momentum dumping requirement (vector) in orbit frame

Δ{right arrow over (H)}_(ECI)=momentum dumping requirement (vector) in Earth—Centered Inertial frame

ΔP_(K) ₁ =spacecraft mass×minimum delta velocity required to control mean K₁

ΔP_(H) ₁ =spacecraft mass×minimum delta velocity required to control mean H₁

ΔP_(Drift)=spacecraft mass×minimum delta velocity required to control mean Drift

{right arrow over (R)}_(i)=lever arm (vector) about the c.g. for the i^(th) thruster in spacecraft body frame {right arrow over (F)}_(i)=thrust vector for the i^(th) thruster in spacecraft body frame

Δt_(i)=on time for the i^(th) thruster

λ_(Eccentricity)=location of the maneuver

C_(Orbit to ECI)=transformation matrix from orbit to ECI frame,

-   -   rotation matrix about the Z by λ_(Eccentricity)

C_(Body to Orbit)=transformation matrix from spacecraft body to orbit frame

{right arrow over (r)}_(i)=C_(Body to Orbit) {right arrow over (R)}_(i)

${\overset{\rightharpoonup}{f}}_{i} = {{C_{{Body}\mspace{14mu} {to}\mspace{14mu} {Orbit}}{\overset{\rightharpoonup}{F}}_{i}} = \begin{bmatrix} f_{i}^{tangential} \\ f_{i}^{radial} \\ f_{i}^{normal} \end{bmatrix}}$

The solution for the two-maneuvers eccentricity control can be used in conjunction with the equation for momentum and drift control to obtain the complete solution for momentum dumping and two maneuvers drift/eccentricity control:

$\mspace{79mu} {{\sum\limits_{{j = 1},2}\; {{\overset{\_}{f}}_{j}^{radial}\Delta \; {\overset{\_}{t}}_{j}}} = {\sum\limits_{{j = 1},2}P_{j}^{radial}}}$ $\mspace{79mu} {{\sum\limits_{{j = 1},2}\; {{\overset{\_}{f}}_{j}^{tangential}\Delta \; {\overset{\_}{t}}_{j}}} = {{\sum\limits_{{j = 1},2}P_{j}^{tangential}} = {{{\Delta \; {P_{drift}\left( {{2\; P_{1}^{tangential}\cos \; \lambda_{1}} + {P_{1}^{radial}\sin \; \lambda_{1}}} \right)}} + \left( {{2\; P_{2}^{tangential}{\cos \left( {\lambda_{1} - {\Delta\lambda}} \right)}} + {P_{2}^{radial}{\sin \left( {\lambda_{1} - {\Delta\lambda}} \right)}}} \right)} = {{{\Delta \; {P_{K_{1}}\left( {{2\; P_{1}^{tangential}\sin \; \lambda_{1}} - {P_{1}^{radial}\cos \; \lambda_{1}}} \right)}} + \left( {{2\; P_{2}^{tangential}{\sin \left( {\lambda_{1} - {\Delta\lambda}} \right)}} - {P_{2}^{radial}{\cos \left( {\lambda_{1} - {\Delta\lambda}} \right)}}} \right)} = {{{\Delta \; P_{H_{1}}} - {2\; P_{1}^{radial}P_{2}^{radial}\sin \; {\Delta\lambda}} - {4\; P_{1}^{tangential}P_{2}^{radial}\cos \; {\Delta\lambda}} - {8\; P_{1}^{tangential}P_{2}^{tangential}\sin \; {\Delta\lambda}} + {4\; P_{1}^{radial}P_{2}^{tangential}\cos \; {\Delta\lambda}}} = 0}}}}}$      λ₂ = λ₁ − Δλ $\mspace{79mu} {{\Delta {\overset{\rightharpoonup}{H}}_{ECI}} = {\sum\limits_{j}{\Delta \; {\overset{\rightharpoonup}{H}}_{{ECI},j}}}}$ $\mspace{79mu} {{\Delta \; {\overset{\rightharpoonup}{H}}_{j}} = {{C_{{Orbit}\mspace{14mu} {to}\mspace{14mu} {ECI}}^{- 1}\left( \lambda_{j} \right)}\Delta \; {\overset{\rightharpoonup}{H}}_{{ECI},j}}}$ $\mspace{79mu} {{\sum\limits_{i}{f_{i,j}^{tangential}\Delta \; t_{i,j}}} = P_{j}^{tangential}}$ $\mspace{79mu} {{\sum\limits_{i}{{{\overset{\rightharpoonup}{r}}_{i,j} \otimes {\overset{\rightharpoonup}{f}}_{i,j}}\Delta \; t_{i,j}}} = {\Delta \; {\overset{\rightharpoonup}{H}}_{j}}}$ $\mspace{79mu} {{\overset{\rightharpoonup}{r}}_{i,j} = {C_{{Body}\mspace{14mu} {to}\mspace{14mu} {Orbit}}{\overset{\rightharpoonup}{R}}_{i,j}}}$ $\mspace{79mu} {{\overset{\rightharpoonup}{f}}_{i,j} = {{C_{{Body}\mspace{14mu} {to}\mspace{14mu} {Orbit}}{\overset{\rightharpoonup}{F}}_{i,j}} = \begin{bmatrix} f_{i,j}^{tangential} \\ f_{i,j}^{radial} \\ f_{i,j}^{normal} \end{bmatrix}}}$      j = 1, 2  index  for  the  maneuvers      i = index  for  the  i^(th)  thruster

The four sets of equations above (momentum dumping and inclination control; momentum dumping and drift control; one maneuver drift and eccentricity control; and two maneuvers drift and eccentricity control) can be performed independently, or in various combinations with one another. Example combinations include momentum dumping and inclination control with one maneuver drift and eccentricity control, and momentum dumping and inclination control with two maneuvers drift and eccentricity control. Under certain circumstances, momentum dumping and drift control may be performed independently in order to maintain the satellite's longitude. For orbits that do not require control of inclination, such as, for example, satellites designed for geo-mobile communications, either one maneuver drift and eccentricity control or two maneuvers drift and eccentricity control may be used to control the orbit drift and eccentricity.

Using the equations described above for simultaneous momentum dumping and orbit control, substantial benefits can be achieved. For example, the number of maneuvers needed to maintain station can be reduced. Also, station-keeping maneuvers can be performed with a single burn. Each of these benefits contributes to increased efficiency in propellant usage, which in turn extends the satellite's lifespan. If desired, single station-keeping maneuvers can be broken into segments, or pulses, which can be spaced out over multiple burns. In such embodiments, the pulses can be separated by lesser time intervals as compared to prior art methods. For example, the elapsed time between pulses may be on the order of minutes, rather than hours, and may even be less than one minute.

The present system and methods also enable tighter orbit control, which has the added benefit of reducing the antenna pointing budget. Because station-keeping maneuvers can be performed with single burns, or with closely spaced pulsed burns, transients are reduced. The satellite is thus more likely to be on station, even between pulses. Station-keeping maneuvers can also be performed with a reduced number of station-keeping thrusters aboard the satellite. For example, some maneuvers can be performed with as little as three or four thrusters.

The present methods also eliminate the need for the thrusters to point through the center of mass of the satellite, which in turn reduces the need for dedicated station-keeping thrusters. In certain embodiments, however, some thrusters may point through the center of mass. The present methods can also be performed with thrusters that are not pivotable with respect to the satellite, which reduces the complexity and cost of the satellite. In certain embodiments, however, some or all thrusters may be pivotable with respect to the satellite. For example, the thrusters may be mounted on gimbaled platforms.

The present system and methods of simultaneous momentum dumping and orbit control also facilitate completely autonomous orbit and ACS control. Satellites are typically controlled from Earth, with station-keeping commands transmitted from Earth to the satellite.

The present methods, however, facilitate elimination of the Earth-bound control center. The satellite itself may monitor its position and trajectory, generate station-keeping commands on board, and execute the commands, all without the need for any intervention from Earth.

While the system and methods above have been described as having utility with geosynchronous satellites, those of ordinary skill in the art will appreciate that the present system and methods may also be used for orbit control and momentum dumping in satellites in non-geosynchronous circular and near circular orbits. For example, the present system and methods may also be used for satellites in non-geosynchronous low Earth orbit (altitude from approximately 100 km to approximately 2,000 km) and/or medium Earth orbit (altitude from approximately 3,000 km to approximately 25,000+km).

The above description presents the best mode contemplated for carrying out the present system and methods for simultaneous momentum dumping and orbit control, and of the manner and process of making and using them, in such full, clear, concise, and exact terms as to enable any person skilled in the art to which they pertain to make this system and use these methods. This system and these methods are, however, susceptible to modifications and alternate constructions from those discussed above that are fully equivalent. Consequently, this system and these methods are not limited to the particular embodiments disclosed. On the contrary, this system and these methods cover all modifications and alternate constructions coming within the spirit and scope of the system and methods as generally expressed by the following claims, which particularly point out and distinctly claim the subject matter of the system and methods. 

1-18. (canceled)
 19. A method of simultaneous orbit control and momentum dumping in a spacecraft, the spacecraft including a plurality of thrusters, the method comprising the steps of: generating a set of firing commands for the thrusters from solutions to momentum dumping and drift control equations; and firing the thrusters according to the firing commands; wherein the momentum dumping and drift control equations are defined as ${\Delta \; \overset{\rightharpoonup}{H}} = {\sum\limits_{i}{{{\overset{\rightharpoonup}{r}}_{i} \otimes {\overset{\rightharpoonup}{f}}_{i}}\Delta \; t_{i}}}$ ${{\sum\limits_{i}{f_{i}^{tangential}\Delta \; t_{i}}} = {\Delta \; P_{Drift}}};$ where Δ{right arrow over (H)}=momentum dumping requirement (vector) in orbit frame ΔP_(Drift)=spacecraft mass×minimum delta velocity required to control mean Drift {right arrow over (R)}_(i)=lever arm (vector) about the c.g. for the i^(th) thruster in spacecraft body frame {right arrow over (F)}_(i)=thrust vector for the i^(th) thruster in spacecraft body frame Δt_(i)=on time for the i^(th) thruster C_(Orbit to ECI)=transformation matrix from orbit to ECI frame C_(Body to Orbit)=transformation matrix from spacecraft body to orbit frame {right arrow over (r)}_(i)=C_(Body to Orbit) {right arrow over (R)}_(i) $\mspace{11mu} {{\overset{\rightharpoonup}{f}}_{i} = {{C_{{Body}\mspace{14mu} {to}\mspace{14mu} {Orbit}}{\overset{\rightharpoonup}{F}}_{i}} = {\begin{bmatrix} f_{i}^{tangential} \\ f_{i}^{radial} \\ f_{i}^{normal} \end{bmatrix}.}}}$
 20. The method of claim 19, wherein the thrusters have fixed orientations relative to the spacecraft, such that the thrusters cannot pivot with respect to the spacecraft.
 21. The method of claim 19, wherein the firing commands generate only a single burn in the thrusters.
 22. The method of claim 19, wherein when each thruster is fired it applies a force to the spacecraft, and none of said forces points through the center of mass of the spacecraft.
 23. The method of claim 19, wherein the thrusters are chemical thrusters or ion thrusters.
 24. The method of claim 19, wherein the firing commands are a first set of firing commands, and further comprising the step of: generating a second set of firing commands for the thrusters from solutions to momentum dumping/drift and eccentricity control equations, wherein the momentum dumping/drift and eccentricity control equations are defined as $P^{tangential} = {\sum\limits_{i}{f_{i}^{tangential}\Delta \; t_{i}}}$ $P^{radial} = {\sum\limits_{i}{f_{i}^{tangential}\Delta \; t_{i}}}$ $\lambda_{Eccentricity} = {\tan^{- 1}\left( \frac{{2\; P^{tangential}\Delta \; P_{H_{1}}} + {P^{radial}\Delta \; V_{K_{1}}}}{{2\; P^{tangential}\Delta \; P_{K_{1}}} - {P^{radial}\Delta \; V_{H_{1}}}} \right)}$ ${\Delta \; {\overset{\rightharpoonup}{H}}_{ECI}} = {C_{{Orbit}\mspace{14mu} {to}\mspace{14mu} {ECI}}\Delta \; \overset{\rightharpoonup}{H}}$ ${\Delta \; \overset{\rightharpoonup}{H}} = {\sum\limits_{i}{{{\overset{\rightharpoonup}{r}}_{i} \otimes {\overset{\rightharpoonup}{f}}_{i}}\Delta \; t_{i}}}$ ${{\sum\limits_{i}{f_{i}^{tangential}\Delta \; t_{i}}} = {\Delta \; P_{Drift}}};$ where Δ{right arrow over (H)}=momentum dumping requirement (vector) in orbit frame Δ{right arrow over (H)}_(ECI)=momentum dumping requirement (vector) in Earth—Centered Inertial frame ΔP_(K) ₁ =spacecraft mass×minimum delta velocity required to control mean K₁ ΔP_(H) ₁ =spacecraft mass×minimum delta velocity required to control mean H₁ ΔP_(Drift)=spacecraft mass×minimum delta velocity required to control mean Drift {right arrow over (R)}_(i)=lever arm (vector) about the c.g. for the i^(th) thruster in spacecraft body frame {right arrow over (F)}_(i)=thrust vector for the i^(th) thruster in spacecraft body frame Δt_(i)=on time for the i^(th) thruster λ_(Eccentricity)=location of the maneuver C_(Orbit to ECI)=transformation matrix from orbit to ECI frame, rotation matrix about the Z by λ_(Eccentricity) C_(Body to Orbit)=transformation matrix from spacecraft body to orbit frame {right arrow over (r)}_(i)=C_(Body to Orbit) {right arrow over (R)}_(i) $\mspace{11mu} {{\overset{\rightharpoonup}{f}}_{i} = {{C_{{Body}\mspace{14mu} {to}\mspace{14mu} {Orbit}}{\overset{\rightharpoonup}{F}}_{i}} = {\begin{bmatrix} f_{i}^{tangential} \\ f_{i}^{radial} \\ f_{i}^{normal} \end{bmatrix}.}}}$
 25. The method of claim 24, wherein the thrusters are fired according to the first and second sets of firing commands simultaneously.
 26. The method of claim 19, wherein the firing commands are a first set of firing commands, and further comprising the step of: generating a second set of firing commands for the thrusters from solutions to momentum dumping/drift and eccentricity control equations wherein the momentum dumping/drift and eccentricity control equations are defined as $\mspace{79mu} {{\sum\limits_{{j = 1},2}\; P_{j}^{tangential}} = {{{\Delta \; {P_{drift}\left( {{2\; P_{1}^{tangential}\cos \; \lambda_{1}} + {P_{1}^{radial}\sin \; \lambda_{1}}} \right)}} + \left( {{2\; P_{2}^{tangential}{\cos \left( {\lambda_{1} - {\Delta\lambda}} \right)}} + {P_{2}^{radial}{\sin \left( {\lambda_{1} - {\Delta\lambda}} \right)}}} \right)} = {{{\Delta \; {P_{K_{1}}\left( {{2\; P_{1}^{tangential}\sin \; \lambda_{1}} - {P_{1}^{radial}\cos \; \lambda_{1}}} \right)}} + \left( {{2\; P_{2}^{tangential}{\sin \left( {\lambda_{1} - {\Delta\lambda}} \right)}} - {P_{2}^{radial}{\cos \left( {\lambda_{1} - {\Delta\lambda}} \right)}}} \right)} = {{{\Delta \; P_{H_{1}}} - {2\; P_{1}^{radial}P_{2}^{radial}\sin \; {\Delta\lambda}} - {4\; P_{1}^{tangential}P_{2}^{radial}\cos \; {\Delta\lambda}} - {8\; P_{1}^{tangential}P_{2}^{tangential}\sin \; {\Delta\lambda}} + {4\; P_{1}^{radial}P_{2}^{tangential}\cos \; {\Delta\lambda}}} = 0}}}}$       λ₂ = λ₁ − Δλ $\mspace{79mu} {{\Delta {\overset{\rightharpoonup}{H}}_{ECI}} = {{\Delta \; {\overset{\rightharpoonup}{H}}_{{ECI},1}} + {\Delta \; {\overset{\rightharpoonup}{H}}_{{ECI},2}}}}$ $\mspace{79mu} {{\Delta \; {\overset{\rightharpoonup}{H}}_{{ECI},1}} = {{C_{{Orbit}\mspace{14mu} {to}\mspace{14mu} {ECI}}\left( \lambda_{1} \right)}\Delta \; {\overset{\rightharpoonup}{H}}_{1}}}$ $\mspace{79mu} {{\Delta \; {\overset{\rightharpoonup}{H}}_{{ECI},2}} = {{C_{{Orbit}\mspace{14mu} {to}\mspace{14mu} {ECI}}\left( \lambda_{2} \right)}\Delta \; {\overset{\rightharpoonup}{H}}_{2}}}$ $\mspace{79mu} {P_{j}^{radial} = {\sum\limits_{i}{f_{i,j}^{radial}\Delta \; t_{i,j}}}}$ $\mspace{79mu} {P_{j}^{tangential} = {\sum\limits_{i}{f_{i,j}^{tangential}\Delta \; t_{i,j}}}}$ $\mspace{79mu} {{{\Delta \; {\overset{\rightharpoonup}{H}}_{j}} = {\sum\limits_{i}{{{\overset{\rightharpoonup}{r}}_{i,j} \otimes {\overset{\rightharpoonup}{f}}_{i,j}}\Delta \; t_{i,j}}}};}$ where {right arrow over (r)}_(i,j)=C_(Body to Orbit) {right arrow over (R)}_(i,j) ${\overset{\rightharpoonup}{f}}_{i,j} = {{C_{{Body}\mspace{14mu} {to}\mspace{14mu} {Orbit}}{\overset{\rightharpoonup}{F}}_{i,j}} = \begin{bmatrix} f_{i,j}^{tangential} \\ f_{i,j}^{radial} \\ f_{i,j}^{normal} \end{bmatrix}}$ j = 1, 2 i = index  for  the  i^(th)  thruster.
 27. The method of claim 26, wherein the thrusters are fired according to the first and second sets of firing commands simultaneously.
 28. A method of simultaneous orbit control and momentum dumping in a spacecraft, the spacecraft including a plurality of thrusters, the method comprising the steps of: generating a set of firing commands for the thrusters from solutions to momentum dumping/drift and eccentricity control equations; and firing the thrusters according to the firing commands; wherein the momentum dumping/drift and eccentricity control equations are defined as $P^{tangential} = {\sum\limits_{i}{f_{i}^{tangential}\Delta \; t_{i}}}$ $P^{radial} = {\sum\limits_{i}{f_{i}^{radial}\Delta \; t_{i}}}$ $\lambda_{Eccentricity} = {\tan^{- 1}\left( \frac{{2\; P^{tangential}\Delta \; P_{H_{1}}} + {P^{radial}\Delta \; V_{K_{1}}}}{{2\; P^{tangential}\Delta \; P_{K_{1}}} - {P^{radial}\Delta \; V_{H_{1}}}} \right)}$ ${\Delta \; {\overset{\rightharpoonup}{H}}_{ECI}} = {C_{{Orbit}\mspace{14mu} {to}\mspace{14mu} {ECI}}\Delta \; \overset{\rightharpoonup}{H}}$ ${\Delta \; \overset{\rightharpoonup}{H}} = {\sum\limits_{i}{{{\overset{\rightharpoonup}{r}}_{i} \otimes {\overset{\rightharpoonup}{f}}_{i}}\Delta \; t_{i}}}$ ${{\sum\limits_{i}{f_{i}^{tangential}\Delta \; t_{i}}} = {\Delta \; P_{Drift}}};$ where Δ{right arrow over (H)}=momentum dumping requirement (vector) in orbit frame Δ{right arrow over (H)}_(ECI)=momentum dumping requirement (vector) in Earth—Centered Inertial frame ΔP_(K) ₁ =spacecraft mass×minimum delta velocity required to control mean K₁ ΔP_(H) ₁ =spacecraft mass×minimum delta velocity required to control mean H₁ ΔP_(Drift)=spacecraft mass×minimum delta velocity required to control mean Drift {right arrow over (R)}_(i)=lever arm (vector) about the c.g. for the i^(th) thruster in spacecraft body frame {right arrow over (F)}_(i)=thrust vector for the i^(th) thruster in spacecraft body frame Δt_(i)=on time for the i^(th) thruster λ_(Eccentricity)=location of the maneuver C_(Orbit to ECI)=transformation matrix from orbit to ECI frame, rotation matrix about the Z by λ_(Eccentricity) C_(Body to Orbit)=transformation matrix from spacecraft body to orbit frame {right arrow over (r)}_(i)=C_(Body to Orbit) {right arrow over (R)}_(i) ${\overset{\rightharpoonup}{f}}_{i} = {{C_{{Body}\mspace{14mu} {to}\mspace{14mu} {Orbit}}{\overset{\rightharpoonup}{F}}_{i}} = {\begin{bmatrix} f_{i}^{tangential} \\ f_{i}^{radial} \\ f_{i}^{normal} \end{bmatrix}.}}$
 29. A method of simultaneous orbit control and momentum dumping in a spacecraft, the spacecraft including a plurality of thrusters, the method comprising the steps of: generating a set of firing commands for the thrusters from solutions to momentum dumping/drift and eccentricity control equations; and firing the thrusters according to the firing commands; wherein the momentum dumping/drift and eccentricity control equations are defined as $\mspace{79mu} {{\sum\limits_{{j = 1},2}\; P_{j}^{tangential}} = {{{\Delta \; {P_{drift}\left( {{2\; P_{1}^{tangential}\cos \; \lambda_{1}} + {P_{1}^{radial}\sin \; \lambda_{1}}} \right)}} + \left( {{2\; P_{2}^{tangential}{\cos \left( {\lambda_{1} - {\Delta\lambda}} \right)}} + {P_{2}^{radial}{\sin \left( {\lambda_{1} - {\Delta\lambda}} \right)}}} \right)} = {{{\Delta \; {P_{K_{1}}\left( {{2\; P_{1}^{tangential}\sin \; \lambda_{1}} - {P_{1}^{radial}\cos \; \lambda_{1}}} \right)}} + \left( {{2\; P_{2}^{tangential}{\sin \left( {\lambda_{1} - {\Delta\lambda}} \right)}} - {P_{2}^{radial}{\cos \left( {\lambda_{1} - {\Delta\lambda}} \right)}}} \right)} = {{{\Delta \; P_{H_{1}}} - {2\; P_{1}^{radial}P_{2}^{radial}\sin \; {\Delta\lambda}} - {4\; P_{1}^{tangential}P_{2}^{radial}\cos \; {\Delta\lambda}} - {8\; P_{1}^{tangential}P_{2}^{tangential}\sin \; {\Delta\lambda}} + {4\; P_{1}^{radial}P_{2}^{tangential}\cos \; {\Delta\lambda}}} = 0}}}}$       λ₂ = λ₁ − Δλ $\mspace{79mu} {{\Delta {\overset{\rightharpoonup}{H}}_{ECI}} = {{\Delta \; {\overset{\rightharpoonup}{H}}_{{ECI},1}} + {\Delta \; {\overset{\rightharpoonup}{H}}_{{ECI},2}}}}$ $\mspace{79mu} {{\Delta \; {\overset{\rightharpoonup}{H}}_{{ECI},1}} = {{C_{{Orbit}\mspace{14mu} {to}\mspace{14mu} {ECI}}\left( \lambda_{1} \right)}\Delta \; {\overset{\rightharpoonup}{H}}_{1}}}$ $\mspace{79mu} {{\Delta \; {\overset{\rightharpoonup}{H}}_{{ECI},2}} = {{C_{{Orbit}\mspace{14mu} {to}\mspace{14mu} {ECI}}\left( \lambda_{2} \right)}\Delta \; {\overset{\rightharpoonup}{H}}_{2}}}$ $\mspace{79mu} {P_{j}^{radial} = {\sum\limits_{i}{f_{i,j}^{radial}\Delta \; t_{i,j}}}}$ $\mspace{79mu} {P_{j}^{tangential} = {\sum\limits_{i}{f_{i,j}^{tangential}\Delta \; t_{i,j}}}}$ $\mspace{79mu} {{{\Delta \; {\overset{\rightharpoonup}{H}}_{j}} = {\sum\limits_{i}{{{\overset{\rightharpoonup}{r}}_{i,j} \otimes {\overset{\rightharpoonup}{f}}_{i,j}}\Delta \; t_{i,j}}}};}$ where {right arrow over (r)}_(i,j)=C_(Body to Orbit) {right arrow over (R)}_(i,j) ${\overset{\rightharpoonup}{f}}_{i,j} = {{C_{{Body}\mspace{14mu} {to}\mspace{14mu} {Orbit}}{\overset{\rightharpoonup}{F}}_{i,j}} = \begin{bmatrix} f_{i,j}^{tangential} \\ f_{i,j}^{radial} \\ f_{i,j}^{normal} \end{bmatrix}}$ j = 1, 2 i = index  for  the  i^(th)  thruster. 30-31. (canceled)
 32. The method of claim 19, wherein the solution results in either under correction or over correction of the eccentricity perturbation, and wherein the method further comprises: correcting a difference in a next control cycle.
 33. The method of claim 19 further comprising: firing the thrusters according to the firing commands to perform completely autonomous orbit and attitude control system control.
 34. The method of claim 19 further comprising: finding a closed form solution to momentum dumping and drift control equations by coupling momentum dumping with orbit control in specified directions.
 35. The method of claim 19 further comprising: performing a momentum dump.
 36. The method of claim 35 further comprising: performing the momentum dump in conjunction with drift control.
 37. The method of claim 35 further comprising: performing the momentum dump in conjunction with inclination control.
 38. The method of claim 35 further comprising: performing the momentum dump in conjunction with both drift control and inclination control.
 39. The method of claim 19 further comprising: performing the momentum dump in conjunction with eccentricity control.
 40. The method of claim 19 further comprising: performing momentum dumping and drift control independently to maintain a longitude of the spacecraft.
 41. The method of claim 19 further comprising: performing station-keeping maneuvers in pulses spaced out over multiple burns, wherein an elapsed time between the pulses comprises about a second to about minutes. 